Method for measuring fluid flow

ABSTRACT

A method for measuring fluid flow includes generating vortices in a fluid and relating the fluid flow to a first set of fluid parameters to obtain a first relationship, and relating the fluid flow to a second set of fluid parameters to obtain a second relationship. The first and second sets of fluid parameters are monitored. A first flow value is calculated from the first set of monitor fluid parameters and the first relationship. The second relationship is adjusted based on the first flow value. The output value is calculated from the second set of monitored fluid parameters and the adjusted second relationship.

This application is a continuation-in-part of application Ser. No. 08/826,167, filed Mar. 27, 1997, which is hereby incorporated by reference in its entirety, now U.S. Pat. No. 6,170,338. This application relates to applications: VORTEX FLOWMETER WITH SIGNAL PROCESSING, Ser. No. 09/400,503; VORTEX FLOWMETER WITH MEASURED PARAMETER ADJUSTMENT, Ser. No. 09/399,898; and ANCILLARY PROCESS OUTPUTS OF A VORTEX FLOWMETER, Ser. No. 09/399,707, all of which are filed on even date herewith and hereby incorporated by reference in their entirety.

BACKGROUND OF THE INVENTION

The present invention relates to flowmeters such as vortex shedding meters or swirlmeters which are responsive to a fluid flow.

Flowmeters sense the flow of liquids or gasses in conduits and produce a signal indicative of the flow. Under certain circumstances, the presence of an obstacle known alternatively as a shedding bar, bluff body, or vortex generator, in a flow conduit causes periodic vortices in the flow. The frequency of these vortices is directly proportional to the flow velocity in the flowmeter. The shedding vortices produce an alternating differential pressure across the bluff body at the shedding frequency. This differential pressure is converted to an electrical signal by piezoelectric crystals or other differential pressure devices. The magnitude of the differential pressure or electric signal is proportional to ρV², where ρ is the fluid density and V is the fluid velocity. When the ratio of pipe diameter to the size of the bluff body is held constant, the signal magnitude is proportional to ρD²F², where D is the inside diameter of the metering pipe and F is the shedding frequency. The vortex flowmeter produces pulses having a frequency proportional to the flow rate. In a swirlmeter, the fluid whose flow rate is to be measured is forced to assume a swirl component by means of swirl blades, the arrangement being such that the swirling motion is transformed into precessional movement to produce fluidic pulses which are sensed to yield a signal whose frequency is proportional to flow rate. See e.g., U.S. Pat. Nos. 3,616,693 and 3,719,080 which disclose examples of swirlmeters and are hereby incorporated by reference.As used herein, “vortex flowmeter” shall include both vortex shedding meters and swirlmeters.

The vortex flowmeter is a measurement transmitter that is typically mounted in the field of a process control industry installation where power consumption is a concern. The vortex flowmeter can provide a current output representative of the flow rate, where the magnitude of current varies between 4-20 mA on a current loop. It is also desirable for the vortex flowmeter to be powered completely from the current loop so that additional power sources need not be used. Thus, the vortex flowmeter measurement transmitter should be able to operate with less than 4 mA in order for the transmitter to adhere to this process control industry communication standard.

It is known to incorporate a microprocessor into a vortex flowmeter. The microprocessor receives digital representations of the output signal from the vortex sensor and computes desired output quantities based on parameters of the digital representation. For instance, a vortex flowmeter can calculate the mass flow rate through the pipe or conduit. It is desirable to provide the calculated mass flow rate approximately ten times per second. For each new calculation of the mass flow rate, the microprocessor must perform many mathematical steps wherein each mathematical step requires a number of clock cycles, thus limiting the rate at which calculated mass flow rates can be provided. Although it would be desirable to use a more powerful microprocessor, which could perform further calculations to improve accuracy, the microprocessor would require more power than is available from the 4-20 mA industry standard discussed above.

Nevertheless, there is a continuing need for a vortex flowmeter having improved accuracy. However, sacrifices should not be made in the update rate nor should power consumption exceed the power available from the current loop.

SUMMARY OF THE INVENTION

A method for measuring fluid flow includes generating vortices in a fluid and relating the fluid flow to a first set of fluid parameters to obtain a first relationship, and relating the fluid flow to a second set of fluid parameters to obtain a second relationship. The first and second sets of fluid parameters are monitored. A first flow value is calculated from the first set of monitor fluid parameters and the first relationship. The second relationship is adjusted based on the first flow value. The output value is calculated from the second set of monitored fluid parameters and the adjusted second relationship.

BRIEF DESCRIPTION OF THE DRAWINGS

FIG. 1 is a block diagram of a vortex flowmeter in accordance with the present invention.

FIG. 1A is a block diagram of a second embodiment of a vortex flowmeter in accordance with the present invention.

FIG. 2 is a flow chart illustrating operation of the vortex flowmeter of the present invention.

FIGS. 3A and 3B are curves of the compressibility factor as a function of pressure at various temperatures for two fluids.

FIG. 4 is a side elevational view of the vortex flowmeter with portions removed.

FIG. 5 is a sectional view of the vortex flowmeter taken along lines 5—5 of FIG. 4.

FIG. 6 is an enlarged sectional view of a portion of FIG. 4.

FIG. 7 is a sectional view taken along lines 7—7 in FIG. 6.

FIG. 8 is a side elevational view of a second embodiment of the vortex flowmeter with portions removed.

FIG. 9 is a sectional view of the vortex flowmeter taken along lines 9—9 of FIG. 8.

FIG. 10 is a sectional view of a vortex flowmeter with another orientation of a streamlined body.

FIG. 11 is a front elevational view of the vortex flowmeter of FIG. 10 with portions removed.

DETAILED DESCRIPTION OF THE PREFERRED EMBODIMENTS

FIG. 1 illustrates an embodiment of a vortex flowmeter 10 of the present invention. Generally, the vortex flowmeter 10 includes a vortex sensor assembly 11 that includes appropriate mechanical and electrical elements to sense vortices 15 in a fluid 14 that flows through a conduit 16. The vortex sensor 11 is operably coupled to an electronic circuit 12. The electronic circuit 12 produces both a 4-20 mA current on a current loop 17 indicative of flow as well as a square wave output F_(out) having a frequency proportional to fluid flow.

The vortex flowmeter 10 includes a vortex meter housing or flowtube 22 having a vortex generator or bluff body 24 located therein. When the fluid 14 flows past the bluff body FIG. 24, shedding vortices 15 having a frequency indicative of the flow rate are produced. A transducer 26 of the vortex sensor assembly 11, preferably located at the bluff body 24, senses a pressure difference associated with the shedding vortices 15. The vortex sensor 26 can include, for example, a piezoelectric sensor. The sensor 26 has characteristics approximated by a potential source E_(s) and a series capacitor C_(s). The magnitude of the output signal from the piezoelectric sensor 26 is proportional to the differential pressure, which is proportional to ρV², where ρ is the fluid density and V is the velocity of the fluid 14, and also proportional to ρD²F², where D is the inside diameter of the meter housing 22 and F is the shedding frequency of the vortices 15.

The output of the transducer 26 is coupled to an amplifier 28 which includes capacitor C_(F) and a resistor R_(F). The amplifier 28 provides an analog output signal on line 30. The signal on line 30 is provided to input circuitry 60 including an anti-aliasing filter 62 and an analog-digital (sigma-delta) converter indicated at 64. The anti-aliasing filter 62 filters the signal from line 30 to remove unwanted high-frequency noise and performs anti-aliasing filtering.

The analog-digital converter 64 samples the signal from filter 62 at approximately 307.2 kHz and outputs a single bit datastream at 307.2 kHz which is indicative of the amplitude and frequency of the vortices 15. There are no word boundaries in the datastream. The relative number of ones and zeros, sometimes called the bit density, is representative of the signal on line 30. The analog-digital converter 64, which is preferably implemented in a CMOS ASIC to minimize power, cost, and size, is particularly suited to digitizing analog signals in the 1 to 10 kHz range, which is a typical frequency range for vortex flowmeters. The digital datastream is transmitted across an electrical isolation barrier 66 required for sensors which are grounded or have leakage current to ground. Such sensors are typically used in vortex flowmeters to reduce cost and simplify connections. The single bit datastream enables an inexpensive, compact transformer or capacitor to be used in the isolation barrier 66. Other isolation media are acceptable such as optical, piezoelectric/acoustic and magnetostrictive isolation means.

The single bit datastream is provided through the isolation barrier 66 to a digital tracking filter 68. The digital tracking filter 68 minimizes frequency quantization noise present in the analog-digital converter 64, and also converts the amplitude and frequency vortex sensor signal on line 30 into a flowmeter output indicative of mass flow. The digital filter 68 receives a noise-contaminated input signal related to flow having a fundamental frequency varying responsively to flow. The digital filter 68 filters the input signal with high pass (HP) filter characteristics and preset low pass (LP) filters to produce a filtered signal representative of flow. The frequency characteristic of the HP filter is selected from a family of preselected HP filters having different corner frequencies. In a preferred embodiment, multiple HP filters are used. A microprocessor 70 selects appropriate corner frequencies of the digital filter 68 or suitable control is provided in the digital filter 68 to select the corner frequencies. The digital filter 68 provides a signal related to the amplitude of the signal on line 30 and, which is roughly proportional to the density, ρ_(V), of the fluid. The signal ρ_(V), in turn is used to calculate the mass flow rate M. The ρ_(V) signal is preferred over another signal ρV also available from the digital filter 68 because the digital filter 68 has removed more noise from the ρ_(V) signal. U.S. Pat. No. 5,429,001 assigned to the same assignee as the present application, and which is hereby incorporated by reference, describes in detail operation of the digital filter 68 to provide the ρ_(V) signal. U.S. Pat. No. 5,942,696 entitled “RAPID TRANSFER FUNCTION DETERMINATION FOR A TRACKING FILTER”, and which is also hereby incorporated by reference, discloses an alternative digital tracking filter. However, an error of approximately 5% compared to actual fluid density can exist in the ρ_(V) signal obtained from either of these digital tracking filters. This error is attributable to the fluid effects on the bluff body 24.

In one aspect of the present invention, the vortex flowmeter 10 improves the accuracy of the output value indicative of flow rate, typically mass flow rate M, by monitoring additional parameters of the fluid 14 flowing in the conduit 16 and using the additional parameters to calculate the desired output value indicative of the flow rate. In the embodiment illustrated, the temperature and the pressure of the fluid 14 flowing in the conduit 16 are measured and provided as an input 80 to the microprocessor 70 The temperature is measured with a suitable temperature sensor 82 such as an RTD (resistive temperature device) or a thermocouple that senses a temperature of the fluid 14, upstream or downstream from the bluff body 24. In the embodiment illustrated, the temperature sensor 82 is disposed in a streamlined body 84 such as an airfoil for ruggedness and to minimize pressure drop along conduit 16. A suitable pressure sensor 86 senses the line pressure of the fluid in the conduit 16. The temperature sensor 82 and the pressure sensor 86 provide output signals to suitable analog-digital converters indicated at 64 (filtering can be provided if necessary). The analog-digital converters 64 transmit corresponding digital signals across the isolation barrier 66 to a decoder 88 that, in turn, provides the signal 80 to the microprocessor 70. In the embodiment illustrated, both the temperature sensor 82 and the pressure sensor 86 are located downstream from the bluff body 24 to avoid disturbing the generation of vortices 15. In a preferred embodiment, the temperature sensor 82 is located approximately six times the inside diameter of the meter housing 22 from the bluff body 24, while the pressure sensor 86 is located approximately four times the inside diameter of the meter housing 22 from the bluff body 24. At these locations, output values obtained from the temperature sensor 82 and the pressure sensor 86 have negligible errors and can be used to calculate fluid density ρ_(V).

FIG. 2 illustrates a flow chart depicting overall operation of the vortex flowmeter 10. The flow chart begins at step 100. From step 100, program flow can be considered as operating along parallel paths indicated at 101 and 103. In practice, the vortex flowmeter 10 executes operational steps in path 101 and performs successive iterations through path 101 before completing a single iteration through path 103. Specifically, the microprocessor 70 will execute operational steps in path 103 in the “background” wherein these steps, or portions thereof, are completed when time is available during or at the completion of the operational steps of path 101. As will be described below, the operational steps of path 101 provide, as a result, the desired output value indicative of flow, herein the mass flow rate M of the fluid 14 in the conduit 16. However, during normal operation of the vortex flowmeter 10, the accuracy of the calculated mass flow rate M is improved by correcting for temperature and pressure of the fluid 14 through the operational steps of path 103.

Referring first to path 101, at step 105, the vortex flowmeter 10 obtains the frequency and amplitude data from the vortex sensor 11, providing that data to the digital tracking filter 68 as described above. The digital tracking filter 68 then provides, at step 107, the density ρ_(V), which is indicative of the flow of the fluid 14 in the conduit 16. Calculations performed at step 107 include applying a stored scaling constant, β, to account for differences in the sensitivity of the vortex sensor 11 and electronics 12, which can vary from element to element for a given line size, for example, ±30% from nominal. Preferably, β is adjusted such that ρ_(V) substantially corresponds to ρ_(G) or ρ_(L) from step 110 discussed below (i.e. C is approximately equal to one). The density value ρ_(V) is then used by the microprocessor 70 in accordance with known equations to calculate the mass flow rate M (similar to that described in U.S. Pat. No. 5,429,001) at step 109. However, in this embodiment of the vortex flowmeter 10 of the present invention, the density value ρ_(V) is corrected with a calibration factor C that is calculated from the operational steps of path 103. Since the calibration factor C can be dependent upon at least one value of the density ρ_(V), and since the calibration factor C may not have been calculated for the first iteration along path 101, the calibration factor C can be initially set to one.

Referring now to path 103, the microprocessor 70 reads at step 102 fluid parameters, such as temperature and pressure from line 80 and obtains a ρ_(V) that was calculated at 107 and that corresponds in time with the measured temperature and pressure. At this point, program flow will traverse subpaths 103A, 103B, or 103C depending on whether the fluid is a gas or liquid, or whether little or any properties of the fluid is known.

If the fluid is a gas, program flow continues along path 103A. At step 104, the microprocessor 70 calculates a compressibility factor, Z, of the fluid 14 flowing in the conduit 16. There are a number of standards for calculating compressibility factors which have been promulgated by a number of organizations such as the American Gas Association. FIGS. 3A and 3B are representative of the variation in the compressibility factor as a function of pressure at various temperatures for gasses having different constituents. Microprocessor 70 preferably calculates the compressibility factor using stored coefficients associated with a particular fluid. Since one set of coefficients is required for each of a plurality of fluids contemplated, and because the magnitude of the compressibility factor varies significantly, it is preferable to use polynomials of the form: $\frac{1}{Z} = {\sum\limits_{i}{\sum\limits_{j}{A_{ij}\quad \frac{P^{i}}{T^{j}}}}}$

where A_(ij) is a curve fitting derived constant stored in memory (EEPROM) 81, T is the process absolute temperature and P is the absolute pressure, and where i and j preferably take on integer values between 0 and 9, depending on the accuracy required to calculate the compressibility factor. A 63 term polynomial (i=0 to 8, j=0 to 6) suffices for most applications. Polynomials of this form and number of terms reduce the amount of computation over direct calculation methods, thereby reducing the time between updates of the calibration factor C and the operating power requirements of vortex flowmeter 10. Moreover, such a technique obviates a large memory to store many numbers of auxiliary constants, again saving power.

After the compressibility factor, Z, has been calculated at step 104, this value is used at step 106 to calculate a density value ρ_(G) according to the ideal gas law.

If the fluid 14 is a liquid, after step 102, program flow continues along a path 103B. The path 103B includes a step 108 where the density ρ_(L) for the liquid is calculated. The microprocessor 70 preferably calculates ρ_(L) using stored polynomials of the form: $\rho_{L} = {\sum\limits_{k}{\sum\limits_{l}{B_{kl}\quad \frac{P^{k}}{T^{l}}}}}$

where B_(kl) is a curve fitting derived constant stored in memory 81, T is the process absolute temperature and P is the absolute pressure, and where k and l can take on appropriate integer values depending on desired accuracy. If desired, since liquids are substantially incompressible, the term P^(k) can be omitted.

A calibration factor, C, is calculated at step 110 as a function of ρ_(G) or ρ_(L) and Pρ_(V). The calibration factor, C, can be a simple ratio obtained from these values, or, in the alternative, can be a rolling average or a time weighted average.

Subpath 103C represents calculation of a calibration factor C wherein little, if any, is known of the fluid properties of the fluid flowing through the conduit 16. Generally, the calibration factor can be expressed as:

C=C _(ref) +ΔC

where C_(ref) is an average value of the calibration factor and wherein ΔC is a small value calculated as a function of available parameters such as the pressure from the pressure sensor 86, the temperature as measured from the temperature sensor 82, ρ_(V) as calculated at step 107, or any other known parameters of the fluid, for example, the dynamic viscosity. For instance, the microprocessor 70 can calculate a calibration factor for changes of the vortex sensor assembly 11 output in stiffness or elasticity as a function of pressure and temperature. In a further embodiment, the microprocessor 70 can calculate a Reynold's Number using ρ_(V), the velocity of the flowing fluid V (obtained from the shedding frequency), the diameter of the meter and the dynamic viscosity μ, which is a function of temperature and fluid type. Although calculation of the Reynold's Number requires knowing the dynamic viscosity of the fluid, an approximation can be used. The dynamic viscosity can simply be a constant (ignoring any temperature effects) or can also be as a function of temperature of the form: $\frac{1}{\mu} = {\sum\limits_{n}\quad \frac{D_{n}}{T^{n}}}$

depending on the extent of knowledge of the fluid properties wherein D_(n) is curve fitting derived constant, T is the process absolute temperature and n can take on an appropriate integer value, depending on desired accuracy. Knowing the Reynold's Number, the microprocessor 70 can correct the “K Factor” and/or a coefficient of pressure on the bluff body 24 that determines differential pressure (ΔP=C_(P)ρV²). If desired, the microprocessor 70 calculates the calibration factor C using stored polynomials of the form: $C = {\sum\limits_{r}{\sum\limits_{s}{C_{rs}\quad \Delta \quad P^{r}\Delta \quad T^{s}}}}$

where C_(rs) is a curve fitting derived constant stored in memory 81, ΔT is the difference between the actual temperature from a reference temperature and ΔP is the difference between the actual pressure and a reference pressure, and where r and s can take on appropriate integer values, depending on desired accuracy. If desired, values for ρ_(V), μ, mach number or other known characteristics or measured fluid parameters can also be incorporated in this equation.

Once the calibration factor C has been calculated it is then used in step 109 for successive iterations of path 101 until a new calibration factor is again calculated in the background during the successive iterations. The microprocessor 70 provides the final output value to a digital-analog converter 83 for converting the digital value to a 4-20 mA current representative of the flow. A digital communications circuit 85 also can receive the final output value for transmission on the current loop 17 using known formats. If desired, a generator 87 can also receive the final output value of mass flow and through an isolator 89 provide a frequency output F_(out) from a pulse circuit 95. Otherwise, the generator 87 can receive a signal 79 indicative of volumetric flow from the digital tracking filter 68. The microprocessor 70 provides suitable scaling constants to the generator 87 when F_(out) is indicative of volumetric flow. A display 73 provides a user interface for the vortex flowmeter 10.

In this manner, the single microprocessor 70 can be used for all processing thereby minimizing the power consumed by the vortex flowmeter 10, allowing it to be completely powered from the current loop 17. Although steps in path 103 require additional processor time, these calculations can be performed by the microprocessor 70, while still providing the desired update rate for the mass flow rate M. This would not be possible if the microprocessor 70 had to calculate the mass flow signal M solely from the density value ρ_(L) or ρ_(G). Under those circumstances, either the update rate of the microprocessor 70 would have to be reduced to stay within available power limits from the current loop 17, or additional power would have to be provided. In the preferred embodiment, the update rate is maintained without exceeding the available power budget because steps in path 103 are performed at a rate less than the update rate of the mass flow rate M.

FIG. 1A illustrates an exemplary embodiment having two microprocessors 70A and 70B. The microprocessor 70A calculates the mass flow rate M pursuant to the flow chart of FIG. 2 as described above. The microprocessor 70B communicates with the microprocessor 70A through a data bus 71. The microprocessor 70B controls the generator 87 and the display 73, and communicates over the current loop 17 with a remote location, not shown, through the digital-analog converter 83 and the digital communications circuit 85. FIG. 1A illustrates one embodiment where multiple microprocessors 70A and 70B are used to perform operational tasks. Embodiments having more than two microprocessors, or where the operational tasks have been delegated differently are also within the scope of the present invention.

Another aspect of the present invention includes calculating additional corrections or providing alarms for volumetric as well as mass flow for both liquids and gasses using the measured pressure and/or temperature. For example, temperature compensation for the “K factor” (ratio of vortex shedding frequency to volumetric flow rate) due to thermal expansion of the meter housing 22 can be provided. As an example, if the meter housing 22 is made from stainless steel, temperature compensation for K factor due to thermal expansion is approximately 0.3% /100° F. Flowmeter 10 would store both a nominal K factor and a correction factor based on the thermal expansion coefficient and the measured temperature. The microprocessor 70 would then use both the nominal K factor and the correction factor to calculate output flow value.

Another correction includes calculation of pressure and temperature changes in viscosity of the fluid 14 to determine a Reynold's Number correction to the K factor. This correction is particularly useful for higher viscosity liquids flowing at low flow rates in small conduits. Hence, both a nominal Reynold's Number and a correction factor (based on temperature, pressure, and fluid type) would be stored and used by flowmeter 10.

In yet another embodiment, an alarm is provided when incipient cavitation is present in the vortex sensor 11. Incipient cavitation results when the pressure of the fluid 14 is near or below the vapor pressure of the fluid. The following equation represents the minimal allowable line pressure, P_(L), five diameters downstream from the meter 22:

P _(L) =AΔP+BP _(VAP)

where ΔP equals the upstream to downstream pressure drop across the bluff body 24 (Δρ=C_(X) ρV ², where C_(X) is a proportionability constant), A is a constant associated with a localized minimum pressure point on the bluff body 24, P_(VAP) is the vapor pressure of the fluid 14 stored as an equation or as a table in memory 81, and B is a constant indicating a threshold margin near the vapor pressure. For instance, constant A can have a value approximately equal to 2.9 (at five diameters downstream), while constant B can have a value approximately equal to 1.3. Constants A and B may vary depending on the actual location of the measured pressure. Preferably, the microprocessor 70 performs this calculation when the amplitude signal from vortex sensor 11 drops below expected values. If the microprocessor 70 calculates that the line pressure of fluid 14 is approaching the vapor pressure, an alarm can be provided over line 17 or at the display 73 indicating cavitation. Otherwise, an alarm can be provided indicating an error in the vortex flowmeter 10.

In another embodiment, the microprocessor 70 uses the measured pressure and temperature data to calculate if condensation is occurring in the gasses flowing through the vortex flowmeter 10. In such a situation, the microprocessor 70 can provide an alarm indicating operation in the gas condensation region.

In an embodiment for a steam application, the microprocessor 70 calculates the quality of steam by comparing the density value ρ_(G) from the measured pressure and temperature data to the density value ρ_(V) obtained from amplitude measurements. The microprocessor 70 provides a signal indicative of steam quality over the current loop 17 to the remote location.

In yet another embodiment, microprocessor 70 calculates the dynamic pressure on the bluff body 24 from the density ρ_(L) or ρ_(G) and the fluid flow rate, or such amplitude can be inferred from the output from sensor 11. If the dynamic pressure exceeds a predetermined value dependent on a maximum allowable value beyond which fatigue and/or structural damage can occur to the bluff body 24 or the sensor 11, the microprocessor 70 can provide an alarm signal on line 17.

In a further embodiment, the microprocessor 70 compares the values of ρ_(V) with ρ_(L) or ρ_(G) and provides an alarm if a difference between these values exceeds a preselected threshold to indicate failure or degradation of sensor 11 or electronics 12. In addition, the microprocessor 70 can monitor the signals obtained from the temperature sensor 82 and the pressure sensor 86 to ascertain if the signals are outside of usable ranges. If either of these signals are outside the usable range, the microprocessor 70 can stop calculating the calibration factor because values obtained may be in error. In this situation, the microprocessor 70 can provide an alarm indicating that mass flow is only being calculated via path 101 wherein the calibration factor C has been set to a default value such as one or the last usable value. Likewise, the microprocessor 70 can monitor the ρ_(V) signal from the digital filter 68 and calculate the mass flow based only values of ρ_(G) or ρ_(L) if the signal of ρ_(V) appears to be in error. The microprocessor 70 can provide a different alarm if the values ρ_(G) or ρ_(L) are only being used.

Each of the foregoing calculations would require additional processor time from the microprocessor 70 and may be accomplished only with a slower update rate on the calculated corrections and/or alarms because of the multi-tasking of the microprocessor 70. Generally, these corrections are small and would not need updating faster than a 10 to 20 second rate. If desired, an integer multiply function can be provided in the ASIC to assist in these calculations, particularly if the update rates of the correction calculations exceed 20 to 30 seconds. Also, with the integer multiply function in the ASIC, the pressure and temperature values can be corrected for linearity, zero offsets and temperature offset compensation.

In another embodiment, data from the temperature sensor 82 and the pressure sensor 86 can be used to calibrate a new vortex sensor 11 in the event the vortex sensor 11 needs to be replaced. Specifically, if the vortex sensor 11 is replaced, the microprocessor 70 compares the value of ρ_(V) with either values from ρ_(G) or ρ_(L) and adjusts the scaling constant β in memory 81 that equates ρ_(G) or ρ_(L) to ρ_(V) so that C remains substantially equal to one. The microprocessor 70 has then calibrated the new vortex sensor 11 and operation continues pursuant to FIG. 2.

In an alternative embodiment illustrated in FIGS. 4-7, the temperature sensor 82 and the pressure sensor 86 are mounted to the meter housing 22 between connecting flanges 22A and 22B. The temperature sensor 82 is mounted in the streamlined body 84 located upstream or downstream from the bluff body 24. The streamlined body 84 is also illustrated in FIGS. 6-7 and includes an inner recess 102 for receiving the temperature sensor 82, for example, a type-N thermocouple, mounted therein. The streamlined body 84 mounts to the meter housing 22 and extends through a recess 103. Referring also back to FIG. 4, a signal line 104 connects the temperature sensor 82 to the electronics 12 located in a transmitter housing 106.

In this embodiment, a support tube 108 supports the transmitter housing 106 on the meter housing 22. The pressure sensor 86 is disposed in a connecting module 111 between the support tube 108 and the transmitter housing 106. Fluid pressure is provided to the pressure sensor 86 through a passageway 110A having at least one port 112 opening to the fluid 14 between the flanges 22A and 22B. In the embodiment illustrated, the ports 112 are located in the streamlined body 84. The passageway 110 A includes an inner bore 113 and a tube 115. Preferably, the tube 115 includes a loop 115A for a condensation trap. A valve 117 is provided in the passageway 110A to allow replacement of the pressure sensor 86 in the field.

In yet another embodiment illustrated in FIGS. 8 and 9, the temperature sensor 82 and the pressure sensor 86 are mounted to the meter housing 22 between connecting flanges 22A and 22B. The temperature sensor 82 is mounted in a streamlined body 184 located downstream from the bluff body 24. The streamlined body 184 is also illustrated in FIG. 5 and includes an inner recess 186 for receiving the temperature sensor 82, for example, a type-N thermocouple, mounted therein. Referring also back to FIG. 8, a signal line 188 connects the temperature sensor 82 to the electronics 12 located in a transmitter housing 190.

In this embodiment, a support tube 192 supports the transmitter housing 190 on the meter housing 22. The pressure sensor 86 is disposed in the transmitter housing 190. Fluid pressure is provided to the pressure sensor 86 through a passageway 194 having a port 196 through the meter housing 22 and opening to the fluid 14 between the flanges 22A and 22B. In the embodiment illustrated, the pressure port 196 is positioned proximate the bluff body 24, in the embodiment illustrated upstream thereof.

In the foregoing embodiments, the streamlined bodies 84 and 184 are oriented substantially parallel to the bluff body 24. FIGS. 10 and 11 illustrate another orientation of the streamlined body 184. The streamlined body 184 is oriented such that a longitudinal axis 184A of the streamlined body 184 is non-parallel to a longitudinal axis 24A of the bluff body 24. Non-parallel orientation minimizes forces from the shedding vortices exerted upon the streamlined body 184. The axis 184A is oriented substantially orthogonal to the axis 24A; however, as appreciated by those skilled in the art, other non-parallel orientations can be used. For instance, other embodiments can include orienting the axis 184A relative to the axis 24A to form an acute angle 193 between the axes 184A and 24A. In a further embodiment, the acute angle 193 is in the approximate range of 30 degrees to less than 90 degrees.

It should also be noted that the streamlined body 184 need not be disposed on the diameter of the flowtube 16 (as illustrated) but rather, can be disposed off the diameter of the flowtube 16 as illustrated by dashed lines 195A and 195B by way of example. In addition, one streamlined body design may be used in flowtubes of varying diameters so as to minimize manufacturing costs. Generally, the streamlined body 184 is of sufficient length to dispose the temperature sensor 82 at an immersion depth suitable to obtain an accurate temperature measurement within allowable tolerances. As appreciated by those skilled in the art, the immersion depth is further related to the velocity and density of the fluid and the heat transfer capabilities of the fluid, streamlined body 184 and flowtube 22.

As stated above, the temperature sensor 82 can be disposed upstream from the bluff body 24. FIG. 10 illustrates location of a streamlined body 197 and temperature sensor 82 upstream of the bluff body 24. Upstream location of the temperature sensor 82 can realize a more compact structure in view that the measurement of fluid temperature in the shedding vortices is generally inaccurate. The streamlined body 197 is substantially similar to the streamlined body 184. As described above with respect to the streamlined body 184, the streamlined body 197 can be disposed in a non-parallel orientation with respect to the bluff body 24. In this manner, potential disturbances of fluid flow are minimized.

The location of ports 112 and temperature sensor 82 in FIGS. 4-7 and 10-11, the port 196 and temperature sensor 82 in FIGS. 8 and 9, and other convenient locations in the meter housing 22 for obtaining the temperature and pressure of the fluid can include corrections due to the dynamic pressure head (proportional to ρV²) and temperature recovery factor:

ΔT=rV ²/2C _(S)

where C_(S) is the specific heat at constant pressure and r is a recovery factor). The microprocessor 70 uses the measured pressure and temperature in the meter housing 22, the measured density ρ_(V) and calculated density ρ_(G) or ρ_(L), in appropriate thermodynamic, energy and momentum equations to correct for errors due to measurement locations. For instance, pressure in front of the bluff body 24 is related to the pressure at four diameters downstream from the bluff body 24 by the following equation:

P−P _(4D) =C _(P) ρV ²

where P is the pressure ahead of the bluff body 24, P_(4D) is the pressure four diameters downstream from the bluff body 24, C_(P) is a pressure loss coefficient that varies with Reynold's Number, ρ is the density of the fluid and V is the velocity of the fluid. Measurement locations between the mounting flanges 22A can provide better mechanical arrangements for the meter housing 22, less sensitivity to location errors, less conduction errors on the temperature sensor, reduced interference with vortex shedding frequency, and reduced plugging of pressure ports. In this manner, the vortex flowmeter 10 can be assembled entirely at the factory, reducing the overall size and cost of the flowmeter 10, and making installation easier since additional penetration points in the conduit are not needed.

Although the present invention has been described with reference to preferred embodiments, workers skilled in the art will recognize that changes may be made in form and detail without departing from the spirit and scope of the invention. 

What is claimed is:
 1. A method for calculating an output value representative of a flow rate of a fluid, comprising: generating vortices in the fluid; relating the fluid flow to a first set of fluid parameters to obtain a first relationship; relating the fluid flow to a second set of fluid parameters to obtain a second relationship; monitoring the first and second sets of fluid parameters; calculating a first flow value from the first set of monitored fluid parameters and the first relationship; adjusting the second relationship based on the first flow value; and calculating the output value from the second set of monitored fluid parameters and the adjusted second relationship.
 2. The method of claim 1, wherein calculating the output value includes determining the output value to be representative of a mass flow rate of the fluid.
 3. The method of claim 2, wherein relating the fluid flow to the first set of fluid parameters includes relating the fluid flow to at least one of a pressure and temperature of the fluid.
 4. The method of claim 3, wherein relating fluid flow to a second set of fluid parameters includes relating the fluid flow to a frequency and an amplitude associated with the vortices.
 5. The method of claim 2, further comprising: monitoring the fluid temperature with a streamlined body disposed downstream of vortice generation.
 6. The method of claim 1, wherein after calculating the output value, the elements of monitoring the first and second sets of parameters and calculating the output value are repeated at a first sampling rate.
 7. The method of claim 6, wherein the elements of calculating the first flow value and adjusting the second relationship are repeated at a second sampling rate that is slower than the first sampling rate.
 8. A method for calculating an output value representative of a mass flow rate of a fluid, comprising: generating vortices in the fluid and measuring at least one characteristic of the vortices and measuring a temperature of the fluid; calculating a first flow value from the temperature measurement; calculating a second flow value from the measured characteristic of the vortices; calculating a calibration factor as a function of the first flow value and the second flow value; and calculating an output mass flow rate as a function of the calibration factor and the measured characteristic of the vortices.
 9. The method of claim 8 wherein calculating the first flow value includes calculating a density value of the fluid.
 10. The method of claim 9 wherein calculating the second flow value includes calculating a second density value of the fluid.
 11. The method of claim 8, further comprising: monitoring the fluid temperature with a streamlined body.
 12. The method of claim 8, wherein after calculating the output mass flow rate, the elements of calculating a second flow value and calculating the output mass flow rate are repeated at a first sampling rate.
 13. The method of claim 12, wherein the elements of calculating the first flow value and calculating the calibration factor are repeated at a second sampling rate slower than the first sampling rate.
 14. The method of claim 8 wherein calculating the first flow value includes calculating the first flow value as a function of at least one previous first flow value.
 15. The method of claim 14 wherein calculating the first flow value as a function of the at least one previous first flow value includes calculating a rolling average of the at least one previous first flow value.
 16. The method of claim 14 wherein calculating the first flow value as a function of the at least one previous first flow value includes calculating a time-weighted average of the at least one previous first flow value.
 17. The method of claim 8 and further comprising measuring a pressure of the fluid, and wherein calculating the first flow value includes calculating the first flow value as a function of the pressure measurement.
 18. The method of claim 17 and further comprising calculating a compressibility factor of the fluid, and wherein calculating the calibration factor includes calculating the calibration factor as a function of the compressibility factor.
 19. The method of claim 18 wherein calculating the compressibility factor (Z) includes using polynomials generally of the form: $\frac{1}{Z} = {\sum\limits_{i}{\sum\limits_{j}{A_{ij}\quad \frac{P^{i}}{T^{j}}}}}$

where Aij is a curve fitting derived constant, T is the fluid temperature and P is the fluid pressure, and where i and j take on integer values.
 20. A method for calculating an output value representative of a mass flow rate of a fluid, comprising: generating vortices in the fluid; detecting at least one characteristic of the vortices; calculating a flow value from the characteristic of the vortices; calculating a calibration factor as a function of at least one of a pressure of the fluid, a temperature of the fluid, and the flow value; and calculating an output mass flow rate as a function of the calibration factor and the flow value.
 21. The method of claim 20 wherein calculating the calibration factor includes calculating the calibration factor as a function of a dynamic viscosity of the fluid.
 22. The method of claim 21 wherein calculating the calibration function is a function of the dynamic viscosity of the fluid and the temperature of the fluid.
 23. The method of claim 20 wherein calculating the calibration factor includes calculating the calibration factor as a function of a Reynold's Number of the fluid.
 24. The method of claim 20 and further comprising: calculating a second flow value from the characteristic of the vortices; and calculating a second output mass flow rate as a function of the calibration factor and the second flow value.
 25. The method of claim 20 wherein calculation of the calibration factor relates to thermal expansion of the flowtube.
 26. A method for calculating an output value representative of a mass flow rate of a fluid, comprising: repeatedly generating vortices in the fluid; repeatedly detecting at least one characteristic of the vortices; repeatedly calculating a flow value from the characteristic of the vortices; repeatedly calculating a calibration factor as a function of at least one of a pressure of the fluid, a temperature of the fluid, and the flow value; and repeatedly calculating an output mass flow rate as a function of the calibration factor and the flow value and at a rate faster than repeatedly calculating the calibration factor. 